HIGH-STRENGTH COLD-ROLLED STEEL SHEET HAVING EXCELLENT FORMABILITY AND COLLISION CHARACTERISTICS AND HAVING TENSILE STRENGTH OF 980 MPa OR MORE, AND METHOD FOR PRODUCING SAME

ABSTRACT

A high-strength cold-rolled steel sheet, in which the metal structure at a position of ¼ of the sheet thickness satisfies (1) to (4) below. (1) The area ratio of ferrite is 0% or more and 10% or less, with the balance being a hard phase including quenched martensite and retained austenite and including at least one selected from the group consisting of bainitic ferrite, bainite, and tempered martensite. (2) The volume ratio V γ  of retained austenite is 5% to 30%. (3) The area ratio V MA  of an MA structure in which quenched martensite and retained austenite are combined is 3% to 25%, and the average circle-equivalent diameter of the MA structure is 2.0 μm or less. (4) The ratio V MA /V γ  of the area ratio V MA  of the MA structure to the volume ratio V γ  of the retained austenite is 0.50 to 1.50.

TECHNICAL FIELD

The present invention relates to a high-strength cold-rolled steel sheet having a tensile strength of 980 MPa or more and being excellent in formability and crashworthiness and to a method for producing the same. In further detail, the present invention relates to the high-strength cold-rolled steel sheet described above, a high-strength electrogalvanized steel sheet having an electrogalvanized layer formed on a surface of the high-strength cold-rolled steel sheet, a high-strength hot-dip galvanized steel sheet having a hot-dip galvanized layer formed on a surface of the high-strength cold-rolled steel sheet, and a high-strength hot-dip galvannealed steel sheet having a hot-dip galvannealed layer formed on a surface of the high-strength cold-rolled steel sheet, and to a method for producing the same.

BACKGROUND ART

In order to achieve fuel cost reduction of automobiles, transport aircrafts and the like, h is desired to reduce the weight of the automobiles, transport aircrafts and the like. In order to achieve weight reduction, it is effective, for example, to reduce the sheet thickness by using a high-strength steel sheet. However, when the steel sheet is made to have a higher strength, the steel sheet comes to have poorer ductility and stretch-flangeability. thereby degrading the formability into a product shape.

Also, in steel parts for automobiles, a steel sheet whose surface has been subjected to galvanization such as electrogalvanization (which may hereafter be denoted as EG), hot-dip galvanizing (which may hereafter be denoted as GI), or hot-dip galvannealing (which may hereafter be denoted as GA), which may hereafter be comprehensively referred to as galvanized steel sheet, is often used from the viewpoint of corrosion resistance. In these galvanized steel sheets as well, increase in strength and formability is demanded in the same manner as in the above high-strength steel sheet.

For example, Patent Literature 1 discloses a hot-dip galvannealed steel sheet having a metal structure in which martensite and retained austenite are mixedly present in ferrite and having a tensile strength TS of 490 to 880 MPa by reinforcement of the complex structure thereof, thus having a good press formability.

Also, Patent Literature 2 discloses a high-strength steel sheet being excellent in stretch-flangeability in which the steel sheet structure is made of 10 to 50% of a ferrite phase and 10 to 50% of a tempered martensite phase in a volume fraction, with the balance being a hard phase, and in which the average crystal grain size in the steel sheet structure is 10 μm or less.

In the meantime, it is demanded that the steel parts for automobiles are excellent in crashworthiness which is an ability to efficiently absorb an impact generated when the automobiles come into collision. There is known, for example, Patent Literature 3 as a technique for improving the crashworthiness. Patent Literature 3 discloses a high-strength galvanized steel sheet having a maximum tensile strength of 900 MPa or more and being excellent in collision absorption energy in which a dynamic/static ratio as large as that of a steel sheet of 590 MPa class and a maximum tensile strength of 900 MPa or more are compatible with each other, as well as a method for producing the same. This production method is characterized in that, after performing galvanization, cooling is performed, and rolling is performed with use of a roll having a roughness (Ra) of 3.0 or less.

CITATION LIST Patent Literature

Patent Literature 1: Japanese Patent No. 3527092

Patent Literature 2: Japanese Patent No. 5021108

Patent Literature 3: Japanese Patent No. 5487916

SUMMARY OF INVENTION Problems to be Solved by the Invention

According to the techniques disclosed in Patent Literatures 1 and 2, the formability of a steel sheet can be improved. However, no consideration is made on the crashworthiness. In contrast, according to the technique disclosed in Patent Literature 3, the crashworthiness of the steel sheet can be improved. However, no consideration is made on the formability as evaluated by ductility and stretch-flangeability.

The present invention has been made in view of the aforementioned circumstances, and an object thereof is to provide a high-strength cold-rolled steel sheet having a tensile strength of 980 MPa or more, having good formability as evaluated by ductility and stretch-flangeability, and having excellent crashworthiness. Another object of the present invention is to provide a high-strength electrogalvanized steel sheet having an electrogalvanized layer on a surface of the high-strength cold-rolled steel sheet, a high-strength hot-dip galvanized steel sheet having a hot-dip galvanized layer on a surface of the high-strength cold-rolled steel sheet, and a high-strength hot-dip galvannealed steel sheet having a hot-dip galvannealed layer on a surface of the high-strength cold-rolled steel sheet. Still another object of the present invention is to provide a method for producing a high-strength cold-rolled steel sheet, a high-strength hot-dip galvanized steel sheet, and a high-strength hot-dip galvannealed steel sheet having the above properties in combination.

Means for Solving the Problems

A high-strength cold-rolled steel sheet having a tensile strength of 980 MPa or more according to the present invention that has solved the aforementioned problems is a steel sheet containing, in mass%, C: 0.10% or more to 0.5% or less. Si: 1.0% or more to 3% or less, Mn: 1.5% or more to 7% or less, P: more than 0% to 0.1% or less. S: more than 0% to 0.05% or less, A1: 0.005% or more to 1% or less, N: more than 0% to 0.01% or less, and O: more than 0% to 0.01% or less, with a balance being iron and inevitable impurities. Further, the gist lies in that a metal structure at a position of 1/4 of a sheet thickness satisfies (1) to (4) below. The torn “MA” is an abbreviation for Martensite-Austenite Constituent.

(1) When the metal structure is observed with a scanning electron microscope, an area ratio of ferrite relative to a whole of the metal structure is 0% or more to 10% or less, with a balance being a hard phase including quenched martensite and retained austenite and including at least one selected from the group consisting of bainitic ferrite, bainite, and tempered martensite. (2) When the metal structure is measured by X-ray diffractometry, a volume ratio V_(γ) of retained austenite relative to the whole of the metal structure is 5% or more to 30% or less. (3) When the metal structure is observed with an optical microscope, an area ratio V_(MA) of an MA structure, in which quenched martensite and retained austenite are combined, relative to the whole of the metal structure is 3% or more to 25% or less, and an average circle-equivalent diameter of the MA structure is 2.0 μm or less. (4) A ratio V_(MA)/V_(γ) of the area ratio V_(MA) of the MA structure to the volume ratio V_(γ) of the retained austenite satisfies a formula (i) below:

0.50≦V _(MA) /V _(γ)≦1.50   (i).

The steel sheet may further contain, as other elements, in mass %:

(a) at least one selected from the group consisting of Cr: more than 0% to 1% or less and Mo: more than 0% to 1% or less, (b) at least one selected from the group consisting of 11: more than 0% to 0.15% or less, Nb: more than 0% to 0.15% or less, and V: more than 0% to 0.15% or less. (c) at least one selected from the group consisting of Cu: more than 0% to 1% or less and Ni: more than 0% to 1% or less, (d) B: more than 0% to 0.005% or less, (e) at least one selected from the group consisting of Ca: more than 0% to 0.01% or less, Mg: more than 0% to 0.01% or less, and REM: more than 0% to 0.01% or less, and the like.

A high-strength electrogalvanized steel sheet having an electrogalvanized layer on a surface of the high-strength cold-rolled steel sheet, a high-strength hot-dip galvanized steel sheet having a hot-dip galvanized layer on a surface of the high-strength cold-rolled steel sheet, and a high-strength hot-dip galvannealed steel sheet having a hot-dip galvannealed layer on a surface of the high-strength cold-rolled steel sheet are also comprised within the scope of the present invention.

The high-strength cold-rolled steel sheet having a tensile strength of 980 MPa or more and being excellent in formability and crashworthiness according to the present invention can be produced by subjecting a steel satisfying a component composition described above to hot rolling with a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being the Ar₃ point or higher to 900° C. or lower, coiling with a coiling temperature being 600° C. or lower, and cooling to room temperature; cold rolling; heating, at an average healing rate of 10° C./second or more, to a temperature region of the Ac₃ point or higher, and soaking by holding in the temperature region for 50 seconds or more; cooling at an average cooling rate of 10° C./second or more, to on arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and the Ms point or lower; and heating and holding in a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower for 50 seconds or more, and thereafter cooling to room temperature.

A high-strength hot-dip galvanized steel sheet having a tensile strength of 980 MPa or more and being excellent in formability and crashworthiness according to the present invention can be produced by subjecting a steel satisfying a component composition described above to hot rolling with a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being the Ar₃ point or higher to 900° C. or lower, coiling with a coiling temperature being 600° C. or lower, and cooling to room temperature; cold rolling; heating, at an average heating rate of 10° C./second or more, to a temperature region of the Ac₃ point or higher, and soaking by holding in the temperature region for 50 seconds or more; cooling at an average cooling rate of 10° C./second or more, to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and the Ms point or lower; and heating and holding in a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower for 50 seconds or more, and after performing hot-dip galvanizing within a holding time, cooling to room temperature.

A high-strength hot-dip galvannealed steel sheet having a tensile strength of 980 MPa or more and being excellent in formability and crashworthiness according to the present invention can be produced by subjecting a steel satisfying a component composition described above to hot rolling width a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being the Ar₃ point or higher to 900° C. or lower, coiling with a coiling temperature being 600° C. or lower, and cooling to room temperature; cold rolling; heating, at an average heating rate of 10° C./second or more, to a temperature region of the Ac₃ point or higher, and soaking by holding in the temperature region for 50 seconds or more; cooling at an average cooling rate of 10° C./second or more, to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and the Ms point or lower; and heating and holding in a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower for 50 seconds or more, and after performing hot-dip galvanizing within a holding time, further performing an alloying treatment and thereafter cooling to room temperature.

Effects of the Invention

According to the present invention, the component composition and the metal structure are suitably controlled, so that a high-strength cold-rolled steel sheet, a high-strength electrogalvanized steel sheet, a high-strength hot-dip galvanized steel sheet, and a high-strength hot-dip galvannealed steel sheet having a tensile strength of 980 MPa or more and being excellent both in formability as evaluated by ductility and stretch-flangeability and in crashworthiness can be provided. The high-strength cold-rolled steel sheet, the high-strength electrogalvanized steel sheet, the high-strength hot-dip galvanized steel sheet, and the high-strength hot-dip galvannealed steel sheet according to the present invention is particularly excellent in stretch-flangeability among the formability properties. The present invention can also provide a method for producing the high-strength cold-rolled steel sheet, the high-strength electrogalvanized steel sheet, the high-strength hot-dip galvanized steel sheet, and the high-strength hot-dip galvannealed steel sheet described above. The high-strength cold-rolled steel sheet, the high-strength electrogalvanized steel sheet, the high-strength hot-dip galvanized steel sheet, and the high-strength hot-dip galvannealed steel sheet according to the present invention are extremely useful in the fields of industry such as automobiles.

BRIEF DESCRIPTION OF DRAWINGS

FIG. 1 is a schematic descriptive view showing one example of a heat treatment pattern performed in the Examples.

DESCRIPTION OF EMBODIMENTS

The present inventors have repeatedly made eager studies in order to improve all of ductility, stretch-flangeability, and crashworthiness in a high-strength cold-rolled steel sheet having a tensile strength of 980 MPa or more. As a result, the present inventors have found out that, in order to improve the ductility while ensuring the tensile strength by setting a ferrite fraction in the metal structure to be a predetermined amount or less and setting the balance structure to be a hard phase, it is effective to appropriately control a ratio V_(MA)/V_(γ) of an area ratio V_(MA) of an MA structure, in which quenched martensite and retained austenite are combined, to a volume ratio V_(γ) of retained austenite relative to the whole of the metal structure and that, in order to improve the stretch-flangeability, it is effective to set the ferrite fraction in the metal structure to be a predetermined amount or less and to make the MA structure finer and, in order to improve the crashworthiness, it is effective to make the MA structure finer and to appropriately control the above ratio V_(MA)/V_(γ) thereby completing the present invention.

First, the metal structure characterizing the present invention will be described.

The high-strength cold-rolled steel sheet according to the present invention is characterized in that the metal structure at a position of ¼ of the sheet thickness satisfies (1) to (4) below.

(1) When the metal structure is observed with a scanning electron microscope, the area ratio of ferrite relative to the whole of the metal structure is 0% or more and 10% or less, with the balance being a hard phase including quenched martensite and retained austenite and including at least one selected from the group consisting of bainitic ferrite, bainite, and tempered martensite. (2) When the metal structure is measured by X-ray diffractometry, the volume ratio V_(γ) of retained austenite relative to the whole of the metal structure is 5% or more and 30% or less. (3) When the metal structure is observed with an optical microscope, the area ratio V_(MA) of an MA structure, in which quenched martensite and retained austenite are combined, relative to the whole of the metal structure is 3% or more and 25% or less, and an average circle-equivalent diameter of the MA structure is 2.0 μm or less. (4) The volume ratio VT of the retained austenite and the area ratio V_(MA) of the MA structure satisfy a formula (i) below:

0.50≦V _(MA) /V _(γ)≦1.50   (i).

The observation of the above metal structure is carried out all at the position of ¼ of the sheet thickness, as representing the steel sheet.

Methods of measuring the fractions in the metal structure as defined in the above (1) to (3) may differ from each other, so that a sum of the fractions may exceed 100%. In other words, in the above (1), the metal structure is observed with a scanning electron microscope, so that the measured area ratio is a ratio obtained when the whole of the metal structure is assumed to be 100%. The area ratio measured with use of a scanning electron microscope includes that of quenched martensite and retained austenite as an area ratio of the hard phase. On the other hand, in the above (2), the retained austenite fraction in the metal structure is calculated by X-ray diffractometry, while in the above (3), the area ratio of the MA structure in which quenched martensite and retained austenite are combined is observed with an optical microscope. For this reason, the fraction of retained austenite and quenched martensite is measured in a duplicated manner by a plurality of methods. Accordingly, a sum of the fractions in the metal structure as defined in the above (1) to (3) may exceed 100%. Also, hereafter, the retained austenite may be denoted as retained γ. Further, the structure in which quenched martensite and retained γ are combined may be denoted as MA structure.

(1) In the present invention, the area ratio of ferrite relative to the whole of the metal structure is set to be 0% or more and 10% or less when the metal structure is observed with a scanning electron microscope. The stretch-flangeability can be improved by suppressing the ferrite amount to be 10 area % or less. In other words, since the high-strength cold-rolled steel sheet according to the present invention is mainly made of a hard phase, the strength can be increased. On the other hand, since ferrite is a soft structure, the difference in strength between the ferrite and the hard phase is large. Accordingly, when the ferrite amount increases, the stretch-flangeability decreases. Also, when ferrite is excessively large in amount, the strength of the steel sheet decreases, making it impossible to ensure a tensile strength of 980 MPa or more. Accordingly, the area ratio of ferrite is set to be 10% or less in the present invention. The area ratio of ferrite is preferably 7% or less, more preferably 5% or less. The ferrite amount is preferably as small as possible, and is most preferably 0 area %.

The balance of the above metal structure is a hard phase including quenched martensite and retained γ as an essential structure and including at least one selected from the group consisting of bainitic ferrite, bainite, and tempered martensite. These hard phases constitute a structure that is harder than ferrite, so that, by making the balance structure be a hard phase while suppressing the ferrite amount to be a predetermined value or less, the strength of the steel sheet can be enhanced to be 980 MPa or more. The reason why quenched martensite and retained γ are contained as an essential structure is, as described later, for the purpose of generating a predetermined amount of an MA structure in which quenched martensite and retained γ are combined.

In addition to the hard phase, the above metal structure may contain at least one selected from the group consisting of pearlite and cementite. A sum area ratio of pearlite and cementite is not particularly limited as long as the effect of the present invention is not deteriorated; however, the sum area ratio is preferably, for example, 20% or less. The sum area ratio is more preferably 15% or less, still more preferably 10% or less.

The area ratio of the above metal structure may be calculated by performing observation with a scanning electron microscope after the position of ¼ of the sheet thickness is corroded with nital, and the observation magnification may be set to be, for example, 1000 times.

(2) In the present invention, when the metal structure is measured by X-ray diffractometry, the volume ratio V_(γ) of retained γ relative to the whole of the metal structure is set to be 5% or more to 30% or less. The retained γ produces an effect of suppressing concentration of strain by receiving the strain so as to be deformed and transformed into martensite when the steel sheet is processed, thereby promoting hardening of the deformed portion during the processing. For this reason, the strength-elongation balance of the steel sheet is enhanced, and the ductility can be improved. In order that such an effect may be exhibited, it is necessary that the volume ratio of retained γ is set to be 5% or more. The volume ratio of retained γ is preferably 6% or more, more preferably 7% or more. However, when the volume ratio of retained γ increases excessively, the stretch-flangeability becomes deteriorated. Accordingly, the volume ratio of retained γ is set to be 30% or less in the present invention. The volume ratio of retained γ is preferably 25% or less, more preferably 20% or less.

The above volume ratio of retained γ may be determined by measuring the position of ¼ of the sheet thickness by X-ray diffractometry. The retained γ exists between the laths of bainitic ferrite or by being included in the MA structure. The above effect by the retained γ is exhibited irrespective of the existence form, so that, in the present invention, the volume ratio was determined by calculating a sum of the amounts of all the retained γ measured by X-ray diffractometry irrespective of the existence form.

(3) In the present invention, when the metal structure is observed with an optical microscope, the area ratio V_(MA) of the MA structure relative to the whole of the metal structure is set to be 3% or more to 25% or less. The above MA structure is a structure that enhances the strength-elongation balance of the steel sheet and can improve the ductility. In order that such an effect may be exhibited, it is necessary that the area ratio of the MA structure is set to be 3% or more. The area ratio of the MA structure is preferably 4% or more, more preferably 5% or more. However, when the area ratio of the MA structure increases excessively, the crashworthiness becomes deteriorated. Accordingly, the area ratio of the MA structure is set to be 25% or less in the present invention. The area ratio of the MA structure is preferably 23% or less, more preferably 20% or less.

Also, in the present invention, the average circle-equivalent diameter of the MA structure is set to be 2.0 μm or less. By making the MA structure be finer, the stretch-flangeability and the crashworthiness can be enhanced. In order that such an effect may be exhibited, it is necessary that the average circle-equivalent diameter of the MA structure is set to be 2.0 μm or less. The average circle-equivalent diameter of the MA structure is preferably 1.8 μm or less, more preferably 1.5 μm or less. According as the MA structure becomes finer, the stretch-flangeability and the crashworthiness will be better, so that a lower limit of the average circle-equivalent diameter of the MA structure is not particularly limited; however, from an industrial point of view, the lower limit is about 0.1 μm.

The above MA structure is a structure in which quenched martensite and retained γ are combined. The quenched martensite means a structure in a state in which untransformed austenite is transformed into martensite during the process in which the steel sheet is cooled from the heating temperature down to room temperature. By observation with an optical microscope, the quenched martensite can be distinguished from the tempered martensite that has been tempered by a heating treatment. In other words, when the metal structure is observed with an optical microscope after being subjected to LePera corrosion, the quenched martensite is observed to be white whereas the tempered martensite is observed to be gray.

The quenched martensite and the retained γ are hardly distinguished from each other by observation with an optical microscope, so that the structure in which quenched martensite and retained γ are combined is measured as the MA structure in the present invention.

The area ratio of the above MA structure is a value as measured at the position of ¼ of the sheet thickness of the steel sheet.

The average circle-equivalent diameter of the MA structure is a value determined by calculating a circle-equivalent diameter based on the area of each MA structure for all the MA structures that are recognized in the field of observation and calculating an average of the obtained circle-equivalent diameters.

(4) In the present invention, it is important that the ratio V_(MA)/V_(γ) of the area ratio V_(MA) of the MA structure to the volume ratio V_(γ) of the retained γ satisfies the following formula (i):

0.50≦V _(MA) /V _(γ)≦1.50   (i).

The ductility and the crashworthiness are rendered compatible with each other when the value of the above ratio V_(MA)/V_(γ) is controlled to satisfy the above formula (i). In other words, as described above, the retained γ is positively generated in the present invention in order to enhance the strength-elongation balance that constitutes an index of ductility. As a result of this, the MA structure is inevitably formed in the steel sheet. Further, upon further studies on the strength-elongation balance, it has been found out that, when a predetermined amount of retained γ is generated, it is good to control the area ratio V_(MA) of the MA structure so that the value of the above ratio V_(MA)/V_(γ) may become 0.50 or more. The value of the above ratio V_(MA)/V_(γ) is preferably 0.55 or more, more preferably 0.60 or more. However, when the value of the above ratio V_(MA)/V_(γ) becomes excessively large, the MA structure is excessively generated. The quenched martensite that exists in the MA structure is a very hard structure, so that, when the MA structure is excessively generated, cracks are liable to be generated at the interface to other structures at the time of collision, and accordingly, the crashworthiness is rather deteriorated. Therefore, in the present invention, the value of the above ratio V_(MA)/V_(γ) is set to be 1.50 or less in order to reduce the area ratio of quenched martensite in the MA structure to ensure the crashworthiness. The value of the above ratio V_(MA)/V_(γ) is preferably 1.40 or less, more preferably 1.30 or less.

As shown above, the metal structure of the high-strength cold-rolled steel sheet that characterizes the present invention has been described.

Next, the component composition of the high-strength cold-rolled steel sheet according to the present invention will be described. Hereafter, “%” with regard to the component composition of a steel sheet means “mass %”.

C: 0.10% or More to 0.5% or Less

C is an element that is necessary for ensuring the tensile strength of 980 MPa or more and for enhancing the stability of retained γ to ensure a predetermined amount of the retained γ. In the present invention, the C amount is set to be 0.10% or more. The C amount is preferably 0.12% or more, more preferably 0.15% or more. However, when the C amount is excessively large, the strength after hot rolling increases, so that cracks may be generated during the cold rolling, or the weldability of a final product may decrease. Accordingly, the C amount is set to be 0.5% or less. The C amount is preferably 0.40% or less, more preferably 0.30% or less, and still more preferably 0.25% or less.

Si: 1.0% or More to 3% or Less

Si is an element that acts as a solute-strengthening element and contributes to a higher strength of the steel. Also, Si suppresses generation of carbide and effectively acts for generation of retained γ, so that Si is an element that is necessary for ensuring an excellent strength-elongation balance. In the present invention, the Si amount is set to be 1.0% or more. The Si amount is preferably 1.2% or more, more preferably 1.35% or more, and still more preferably 1.5% or more. However, when the Si amount is excessively large, a considerable scale is formed during the hot rolling to generate scale marks on the surface of the steel sheet, thereby degrading the surface property. Also, the pickling property is degraded as well. Accordingly, the Si amount is set to be 3% or less. The Si amount is preferably 2.8% or less, more preferably 2.6% or less.

Mn: 1.5% or More to 7% or Less

Mn is an element that contributes to a higher strength of the steel sheet by enhancing the hardenability and suppressing the generation of ferrite. Further, Mn is an element that is necessary for stabilizing γ to generate retained γ. In the present invention, the Mn amount is set to be 1.5% or more. The Mn amount is preferably 1.6% or more, more preferably 1.7% or more, still more preferably 1.8% or more, and furthermore preferably 2.0% or more. However, when the Mn amount is excessively large, the strength after hot rolling increases, so that cracks may be generated during the cold rolling, or the weldability of the final product may decrease. Also, when Mn is added in an excessively large amount, Mn is segregated to deteriorate the ductility and the stretch-flangeability. Accordingly, the Mn amount is set to be 7% or less. The Mn amount is preferably 5.0% or less, more preferably 4.0% or less, and still more preferably 3.0% or less.

P: More Than 0% to 0.1% or Less

P is an impurity element that is inevitably contained and, when contained in an excessively large amount, deteriorates the weldability of the final product. Accordingly, the P amount is set to be 0.1% or less in the present invention. The P amount is preferably 0.08% or less, more preferably 0.05% or less. The smaller the P amount is, the better it is. However, it is industrially difficult to set the P amount to be 0%. A lower limit of the P amount is 0.0005% from the industrial point of view.

S: More Than 0% to 0.05% or Less

As with P, S is an impurity clement that is inevitably contained and, when contained in an excessively large amount, deteriorates the weldability of the final product. Also, S forms sulfide-based inclusions in the steel sheet, thereby causing deterioration of the ductility and the stretch-flangeability of the steel sheet. Accordingly, the S amount is set to be 0.05% or less in the present invention. The S amount is preferably 0.01% or less, more preferably 0.005% or less. The smaller the S amount is, the better it is. However, it is industrially difficult to set the S amount to be 0%. A lower limit of the S amount is 0.0001% from the industrial point of view.

Al: 0.005% or More to 1% or Less

Al is an element that acts as a deoxidizer. In order that such an action may be exhibited, the Al amount is set to be 0.005% or more in the present invention. The Al amount is more preferably 0.01% or more. However, when the Al amount is excessively large, the weldability of the final product is considerably deteriorated. Accordingly, the Al amount is set to be 1% or less in the present invention. The Al amount is preferably 0.8% or less, more preferably 0.6% or less.

N: More Than 0% to 0.01% or Less

N is an impurity element that is inevitably contained and, when N is contained in an excessively large amount, nitride is deposited in a large amount to deteriorate the ductility, stretch-flangeability, and crashworthiness. Accordingly, the N amount is set to be 0.01% or less in the present invention. The N amount is preferably 0.008% or less, more preferably 0.005% or less. Since nitride in a small amount contributes to a higher strength of the steel sheet, the N amount may be 0.001% or more.

O: More Than 0% to 0.01% or Less

O is an impurity element that is inevitably contained and, when contained in an excessively large amount, deteriorates the ductility and the crashworthiness. Accordingly, the O amount is set to be 0.01% or less in the present invention. The O amount is preferably 0.005% or less, more preferably 0.003% or less. The smaller the O amount is, the better it is. However, it is industrially difficult to set the O amount to be 0%. A lower limit of the O amount is 0.0001% from the industrial point of view.

The cold-rolled steel sheet according to the present invention satisfies the aforementioned component composition, and the balance is made of iron and inevitable impurities. The inevitable impurities may include the above-mentioned elements such as P, S, N, and O, which may be brought into the steel depending on the circumstances of raw materials, facility materials, production equipment, and the like, and may also include tramp elements such as Pb, Bi, Sb, and Sn.

The cold-rolled steel sheet of the present invention may further contain, as other elements,

(a) at least one selected from the group consisting of Cr more than 0% to 1% or less and Mo: more than 0% to 1% or less, (b) at least one selected from the group consisting of Ti: more than 0% to 0.15% or less, Nb: more than 0% to 0.15% or less, and V: more than 0% to 0.15% or less, (c) at least one selected from the group consisting of Cu: more than 0% to 1% or less and Ni: more than 0% to 1% or less, (d) B: more than 0% to 0.005% or less, (e) at least one selected from the group consisting of Ca: more than 0% to 0.01% or less, Mg: more than 0% to 0.01% or less, and REM: more than 0% to 0.01% or less, and the like.

These elements of (a) to (c) may be contained either alone or in an arbitrary combination. The reason why such ranges have been set is as follows.

(a) At Least One Selected from the Group Consisting of Cr: More Than 0% to 1% or Less and Mo: More Than 0% to 1% or Less

Cr and Mo are each an element that acts to improve the strength of the steel sheet by enhancing hardenability. In order that such an action may be effectively exhibited, the amount of each of Cr and Mo is preferably set to be 0.1% or more, more preferably 0.3% or more. However, when these elements are contained in an excessively large amount, the ductility and the stretch-flangeability decrease. Also excessive addition leads to higher costs. Accordingly, when Cr or Mo is contained alone, the amount is preferably 1% or less, more preferably 0.8% or less, still more preferably 0.5% or less. Cr and Mo may be used either alone or in combination. When Cr and Mo are used in combination, it is preferable that each amount is within the above range of the content when used alone, and a sum of the contents of Cr and Mo is 1.5% or less.

(b) At Least One Selected from the Group Consisting of Ti: More Than 0% to 0.15% or Less, Nb: More Than 0% to 0.15% or Less, and V: More Than 0% to 0.15% or Less

Ti, Nb, and V are each an element that acts to improve the strength of the steel sheet by forming carbide and nitride in the steel sheet and to make prior γ grains finer. In order that such an action may be effectively exhibited, the amount of each of Ti, Nb, and V is preferably set to be 0.005% or more, more preferably 0.010% or more. However, when these elements ore contained in an excessively large amount, carbide is deposited at the grain boundary, so that the stretch-flangeability and the crashworthiness of the steel sheet are deteriorated. Accordingly, in the present invention, the amount of each of Ti, Nb, and V is preferably set to be 0.15% or less, more preferably 0.12% or less, and still more preferably 0.10% or less. These elements may be used either alone or in combination of two or more that are arbitrarily selected.

(c) At Least One Selected from the Group Consisting of Cu: More Than 0% to 1% or Less and Ni: More Than 0% to 1% or Less

Cu and Ni are each an element that acts effectively for generation and stabilization of retained γ. Also, Cu and Ni act to improve the corrosion resistance of the steel sheet. In order that such an action may be effectively exhibited, the amount of each of Cu and Ni is preferably set to be 0.05% or more, more preferably 0.10% or more. However, when Cu is contained in an excessively large amount, the hot formability is deteriorated. Accordingly, when Cu is added alone, the amount of Cu is preferably set to be 1% or less, more preferably 0.8% or less, and still more preferably 0.5% or less. On the other hand, when Ni is contained in an excessively large amount, a higher cost is invited, so that the amount of Ni is preferably set to be 1% or less, more preferably 0.8% or less, and still more preferably 0.5% or less. Cu and Ni may be used either alone or in combination. When Cu and Ni are used in combination, the above action is more likely to be exhibited, and also, by incorporation of Ni, the deterioration of hot formability caused by addition of Cu is more likely to be suppressed. When Cu and Ni are used in combination, a sum of the amounts of Cu and Ni is preferably set to be 1.5% or less, more preferably 1.0% or less.

(d) B: More Than 0% to 0.005% or Less

B is an element that improves hardenability and is an element that acts to allow austenite to exist stably down to room temperature. In order that such an action may be effectively exhibited, the amount of B is preferably set to be 0.0005% or more, more preferably 0.0010% or more, and still more preferably 0.0015% or more. However, when B is contained in an excessively large amount, boride may be generated to deteriorate the ductility. Accordingly, the amount of B is preferably set to be 0.005% or less. The amount of B is more preferably 0.004% or less, still more preferably 0.0035% or less.

(e) At Least One Selected from the Group Consisting of Ca: More Than 0% to 0.01% or Less, Mg: More Than 0% to 0.01% or Less, and REM: More Than 0% to 0.01% or Less

Ca, Mg, and REM are elements that act to finely disperse the inclusions in the steel sheet. In order that such an action may be effectively exhibited, the amount of each of Ca, Mg, and REM is preferably set to be 0.0005% or more, more preferably 0.0010% or more. However, when these elements are added in an excessively large amount, the castability, hot formability, and the like may be deteriorated. Accordingly, the amount of each of Ca, Mg, and REM is preferably set to be 0.01% or less, more preferably 0.008% or less, and still more preferably 0.007% or less. These elements may be used either alone or in combination of two or more that are arbitrarily selected. In the present invention, REM is an abbreviation for Rare earth metal (rare earth element), and is meant to include lanthanoid elements which are fifteen elements from La to Lu, and Sc and Y.

As shown above, the high-strength cold-rolled steel sheet according to the present invention is described.

An electrogalvanized layer, a hot-dip galvanized layer, or a hot-dip galvannealed layer may be formed on a surface of the high-strength cold-rolled steel sheet. In other words, the scope of the present invention includes a high-strength electrogalvanized steel sheet (which may hereafter be referred to as EG steel sheet) having an electrogalvanized layer formed on a surface of the high-strength cold-rolled steel sheet, a high-strength hot-dip galvanized steel sheet (which may hereafter be referred to as GI steel sheet) having a hot-dip galvanized layer formed on a surface of the high-strength cold-rolled steel sheet, and a high-strength hot-dip galvannealed steel sheet (which may hereafter be referred to as GA steel sheet) having a hot-dip galvannealed layer formed on a surface of the high-strength cold-rolled steel sheet.

Next, a method for producing the high-strength cold-rolled steel sheet according to the present invention is described.

The high-strength cold-rolled steel can be produced by subjecting a steel satisfying a component composition described above to hot rolling with a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being the Ar₃ point or higher to 900° C. or lower, coiling with a coiling temperature being 600° C. or lower, and cooling to room temperature; cold rolling; heating, at an average heating rate of 10° C./second or more, to a temperature region of the Ac₃ point or higher, and soaking by holding in the temperature region for 50 seconds or more; cooling at an average cooling rate of 10° C./second or more, to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and the Ms point or lower, and heating and holding in a temperature region of higher than the cooling slop temperature T° C. to 550° C. or lower for 50 seconds or more, and thereafter cooling to room temperature.

Hereafter, the steps will be sequentially described.

Rolling Rate at a Final Stand of Finish Rolling: 5 to 25%

First, a steel satisfying the aforementioned component composition is heated in accordance with a conventional method. A heating temperature is not particularly limited; however, the heating temperature is preferably set to be, for example, 1000 to 1300° C. When the heating temperature is lower than 1000° C., solid solution of carbide is insufficiently formed, and a sufficient strength is hardly obtained. On the other hand, when the heating temperature is higher than 1300° C. the structure of the hot-rolled steel sheet becomes coarse, and also the MA structure of the cold-rolled steel sheet is liable to become coarse. As a result, the crashworthiness lends to decrease.

After the heating, hot rolling is carried out In the present invention, it is important that the rolling rate at a final stand of finish rolling is set to be 5 to 25%. When the rolling rate is less than 5%, the austenite grain size after hoi rolling becomes coarse, and the average circle-equivalent diameter of the MA structure in the cold-rolled steel sheet after annealing becomes large. As a result, the stretch-flangeability decreases. Accordingly, in the present invention, it is necessary that the rolling rate is set to be 5% or more. The rolling rate is preferably 6% or more, more preferably 7% or more, and still more preferably 8% or more. However, when the rolling rate exceeds 25%, the average circle-equivalent diameter of the MA structure also becomes large, leading to deterioration of the stretch-flangeability and crashworthiness. The mechanism therefor is not clear; however, this seems to be because the structure after hot rolling is made non-homogeneous. In the present invention, it is necessary that the rolling rate is set to be 25% or less. The rolling rate is preferably 23% or less, more preferably 20% or less.

Finish Rolling End Temperature: Ar₃ Point or Higher to 900° C. or Lower

When the finish rolling end temperature is lower than the temperature of the Ar₃ point, the steel sheet structure after hot rolling becomes non-homogeneous, and the stretch-flangeability decreases. On the other hand, when the finish rolling end temperature exceeds 900° C., recrystallization of austenite occurs to make the crystal grains become coarse, and the average circle-equivalent diameter of the MA structure in the cold-rolled steel sheet becomes large. As a result, the stretch-flangeability decreases. Accordingly, in the present invention, it is necessary that the finish rolling end temperature is set to be 900° C. or lower. The finish rolling end temperature is preferably 890° C. or lower, more preferably 880° C. or lower.

The temperature of the Ar₃ point was calculated on the basis of the following formula (ii). In the formula, brackets [ ] indicate the content of each element (mass %), and calculation may be made by assuming that the content of an element that is not contained in the steel sheet is 0 mass %.

Ar₃ point (° C.)=910−310×[C]−80×[Mn]−20×[Cu]−15×[Cr]−55×[Ni]−80×[Mo]  (ii)

Coiling Temperature: 600° C. or Lower

When the coiling temperature exceeds 600° C., the crystal grains become coarse, and the average circle-equivalent diameter of the MA structure in the cold-rolled steel sheet becomes large. As a result, the stretch-flangeability decreases. Accordingly, in the present invention, the coiling temperature is set to be 600° C. or lower. The coiling temperature is preferably 580° C. or lower, more preferably 570° C. or lower, and still more preferably 550° C. or lower.

Cold Rolling

After the hot rolling, the steel sheet may be coiled, cooled to room temperature, pickled by a conventional method in accordance with the needs, and subsequently cold-rolled by a conventional method. The cold rolling rate in the cold rolling may be set to be, for example, 30 to 80%.

Annealing

After the cold rolling, annealing is carried out by heating, at an average heating rate of 10° C./sec or more, to a temperature region of the Ac₃ point or higher, and soaking by holding in the temperature region for 50 seconds or more. When the average heating rale of heating to the above temperature region after the cold rolling is lower than 10° C./sec, the austenite grains grow and become coarse during the heating, so that the average circle-equivalent diameter of the MA structure in the cold-rolled steel sheet becomes large, and the stretch-flangeability decreases. Accordingly, in the present invention, the average healing rate is set to be 10° C./sec or more. The average heating rate is preferably 12° C./sec or more, more preferably 15° C./sec or more. An upper limit of the above average heating rate is not particularly limited; however, the average heating rate is typically about 100° C./sec at the maximum.

By setting the soaking temperature to be the Ac₃ point or higher, the generation of ferrite can be suppressed. When the soaking temperature is lower than the temperature of the Ac₃ point, fertile is generated in an excessively large amount, so that the stretch-flangeability cannot be improved. Accordingly, the soaking temperature is set to be the Ac₃ point or higher in the present invention. The soaking temperature is preferably (Ac₃ point+10° C.) or higher, more preferably (Ac₃ point+20° C.) or higher. An upper limit of the soaking temperature is not particularly limited. However, when the soaking temperature is too high, the austenite may be coarsened, so that the soaking temperature is preferably (Ac₃ point+100° C.) or lower, more preferably (Ac₃ point+50° C.) or lower.

When the soaking time is less than 50 seconds, the processed structure remains in the cold-rolled steel sheet, and the ductility is deteriorated. Accordingly, in the present invention, the soaking time is set to be 50 seconds or more. The soaking time is preferably 60 seconds or more. An upper limit of the soaking time is not particularly limited; however, when the soaking time is too long, concentration of Mn into the austenite phase proceeds, and the Ms point may decrease, leading to increase or coarsening of the MA structure. Accordingly, the soaking time is preferably set to be 3600 seconds or less, more preferably 3000 seconds or less.

Regarding the soaking holding in the above temperature region, the steel sheet need not be thermostatically held at the same temperature, so that the steel sheet may be heated and cooled in a fluctuating manner within the above temperature region.

The temperature of the aforementioned Ac₃ point can be calculated on the basis of the following formula (iii) disclosed in “The Physical Metallurgy of Steels” (William C. Leslie, published by Maruzen Co., Ltd. on May 31, 1985, page 273). In the formula, brackets [ ] indicate the content of each element (mass %), and calculation may be made by assuming that the content of an element that is not contained in the steel sheet is 0 mass %.

Ac₃ (° C.)=910−203×[C]^(1/2)−15.2×[Ni]+44.7×[Si]+104×[V]+31.5×[Mo]+13.1×[W]−(30×[Mn]+11×[Cr]+20×[Cu]−700×[P]−400×[Al]−120×[As]−400×[Ti])   (iii)

Cooling

After the above soaking holding, the steel sheet is cooled to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and the Ms point or lower. By cooling down to this temperature range, untransformed austenite can be transformed to martensite and hard bainite phase, and the MA structure also can be made finer. During this period, martensite exists as quenched martensite immediately after the transformation; however, the martensite is tempered while being reheated and held in a later step and remains as tempered martensite. This tempered martensite does not give adverse effects on any of the ductility, stretch-flangeability, and crashworthiness of the steel sheet. However, when the above cooling stop temperature T exceeds the Ms point, martensite is not generated, and the MA structure generated in the reheating holding step at a high temperature becomes coarse, so that the local deformation capability decreases, and the stretch-flangeability cannot be improved. Moreover, because the MA structure is coarsened, the crashworthiness cannot be improved. Accordingly, in the present invention, the cooling stop temperature T is set to be equal to or lower than the temperature of the Ms point. The cooling stop temperature T is preferably (Ms point −20° C.) or lower, more preferably (Ms point −50° C.) or lower. On the other hand, when the cooling stop temperature T is lower than 100° C., retained γ and the MA structure are hardly generated, so that the ductility cannot be improved. Accordingly, in the present invention, a lower limit of the cooling stop temperature T is set to be 100° C. or higher. The cooling stop temperature T is preferably 110° C. or higher, more preferably 120° C. or higher.

The temperature of the aforementioned Ms point can be calculated on the basis of the following formula (iv). In the formula, brackets [ ] indicate the content of each element (mass %), and calculation may be made by assuming that the content of an element that is not contained in the steel sheet is 0 mass %.

Ms point (° C.)=561−474×[C]−33×[Mn]−17×[Ni]−17×[Cr]−21×[Mo]  (iv)

After performing the above soaking and holding, it is important that an average cooling rate down to the cooling stop temperature T that lies in the above temperature range is set to be 10° C./sec or more. Excessive generation of ferrite can be suppressed by appropriately controlling the cooling rate down to the cooling stop temperature T after soaking and holding. In other words, when the average cooling rate is lower than 10° C./sec, ferrite is excessively generated during the cooling, and the stretch-flangeability decreases. Accordingly, in the present invention, the average cooling rate is set to be 10° C./sec or more. The average cooling rate is preferably 15° C./sec or more, more preferably 20° C./sec or more. An upper limit of the above average cooling rate is not particularly limited, and the steel sheet may be cooled by cooling with water or cooling with oil.

Reheating Step

After the steel sheet is cooled down to an arbitrary cooling stop temperature T° C. that lies in the temperature range of 100° C. or higher and the Ms point or lower, it is important that the steel sheet is reheated to a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower, and the steel sheet is held in this temperature region for 50 seconds or more. By reheating to the temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower, the hard phase such as martensite can be tempered, and untransformed austenite can be transformed to bainitic ferrite or bainite. When the reheating is not carried out, the balance between the amounts of generation of retained γ and the MA structure becomes degraded, and the ratio V_(MA)/V_(γ) of the area ratio V_(MA) of the MA structure to the volume ratio V_(γ) of the retained γ cannot be controlled to be within an appropriate range. As a result, the crashworthiness cannot be improved. Further, the hard phase cannot be tempered, and dislocation at a high density is generated. Accordingly, in the present invention, the steel sheet is reheated to a temperature exceeding the cooling stop temperature T after the steel sheet is cooled to the cooling stop temperature T. The reheating temperature is preferably (T+20° C.) or higher, more preferably (T+30° C.) or higher, and still more preferably (T+50° C. or higher. However, when the reheating temperature exceeds 550° C., retained γ and the MA structure are generated only in a slight amount, so that the tensile strength decreases. Accordingly, in the present invention, the reheating temperature is set to be 550° C. or lower. The reheating temperature is preferably 520° C. or lower, more preferably 500° C. or lower, and still more preferably 450° C. or lower.

In the present invention, “reheating” means, as it is stated, healing, that is, raising the temperature from the above cooling stop temperature T. Accordingly, the reheating temperature is a temperature higher than the above cooling stop temperature T. Therefore, even if the reheating temperature is, for example, within a temperature region of 100° C. or higher and 550° C. or lower, this does not fall under the category of the reheating of the present invention if the cooling stop temperature T and the reheating temperature are the same as each other or if the reheating temperature is lower than the cooling stop temperature T.

After the steel sheet is reheated to the temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower, the steel sheet is held in the temperature region for 50 seconds or more. When the reheating holding time is less than 50 seconds, the MA structure is excessively generated, and the ductility cannot be improved. Further, the MA structure becomes coarse, and the average circle-equivalent diameter cannot be appropriately controlled, so that the stretch-flangeability cannot be improved either. Also, the ratio V_(MA)/V_(γ) of the area ratio V_(MA) of the MA structure to the volume ratio V_(γ) of the retained γ cannot be appropriately controlled, so that the crashworthiness cannot be improved either. Furthermore, the hard phase cannot be sufficiently tempered, and also the transformation of untransformed austenite to bainitic ferrite or bainite docs not proceed sufficiently. Accordingly, in the present invention, the reheating holding lime is set to be 50 seconds or more. The reheating holding time is preferably 80 seconds or more, more preferably 100 seconds or more, and still more preferably 200 seconds or more. An upper limit of the reheating holding time is not particularly limited. However, when the holding time is long, the productivity decreases, and the tensile strength lends to decrease. From such viewpoints, the reheating holding time is preferably set to be 1500 seconds or less, more preferably 1000 seconds or less.

After the steel sheet is reheated and held, the steel sheet is cooled to room temperature. An average cooling rate during the cooling is not particularly limited; however, the average cooling rate is preferably, for example, 0.1° C./sec or more, more preferably 0.4° C./sec or more. Further, the average cooling rate is preferably, for example, 200° C./sec or less, more preferably 150° C./sec or less.

Plating Treatment

After the reheating holding, the high-strength cold-rolled steel sheet according to the present invention obtained by cooling to room temperature may be subjected to electrogalvanization, hot-dip galvanizing, or hot-dip galvannealing in accordance with a conventional method.

The electrogalvanization may be carried out, for example, by subjecting the above high-strength cold-rolled steel sheet to energization while immersing the steel sheet into a zinc solution of 50 to 60° C. (particularly 55° C.) so as to perform an electrogalvanization treatment. The plating adhesion amount is not particularly limited and may be. for example, about 10 to 100 g/m² per one surface.

The hot-dip galvanizing may be carried out, for example, by immersing the above high-strength cold-rolled steel sheet into a hot-dip galvanizing bath of 300° C. or higher and 550° C. or lower, so as to perform a hot-dip galvanizing treatment. The plating time may be suitably adjusted so that a desired plating adhesion amount can be ensured. The plating time is preferably set to be, for example, 1 to 10 seconds.

The hot-dip galvannealing may be carried out by performing an alloying treatment after the above hot-dip galvanizing. The alloying treatment temperature is not particularly limited; however, when the alloying treatment temperature is too low, the alloying does not proceed sufficiently, so that the alloying treatment temperature is preferably 450° C. or higher, more preferably 460° C. or higher, and still more preferably 480° C. or higher. However, when the alloying treatment temperature is too high, the alloying proceeds loo much, and the Fe concentration in the plating layer becomes high, thereby deteriorating the plating adhesion property. From such a viewpoint, the alloying treatment temperature is preferably 550° C. or lower, more preferably 540° C. or lower, and still more preferably 530° C. or lower. The alloying treatment time is not particularly limited and may be adjusted so that the hot-dip galvanized layer may be alloyed. The alloying treatment time is preferably, for example, 10 to 60 seconds.

A high-strength hot-dip galvanized steel sheet having a tensile strength of 980 MPa or more and being excellent in formability and crashworthiness according to the present invention can also be produced by subjecting a steel satisfying a component composition described above to hot rolling with a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being the Ar₃ point or higher and 900° C. or lower, coiling with a coiling temperature being 600° C. or lower, and cooling to room temperature; cold rolling; heating, at an average heating rate of 10° C./second or more, to a temperature region of the Ac₃ point or higher, and soaking by holding in the temperature region for 50 seconds or more; cooling at an average cooling rate of 10° C./second or more, to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and the Ms point or lower; and heating and holding in a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower for 50 seconds or more, and after performing hot-dip galvanizing within a holding time, cooling to room temperature. In other words, the steps until heating to the temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower are the same as those of the above-described method for producing a high-strength cold-rolled steel sheet according to the present invention, so that the hot-dip galvanizing and the holding for 50 seconds or more that is carried out in the above temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower may be simultaneously carried out in the same step.

The hot-dip galvanizing may be carried out within the holding time in the reheating temperature region, that is, in the temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower, and a conventional method can be adopted as a specific plating method. For example, the steel sheet heated to the temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower may be immersed into a plating bath adjusted to have a temperature within the range of higher than the cooling stop temperature T° C. to 550° C. or lower, so as to perform a hot-dip galvanizing treatment. The plating time may be suitably adjusted so that a desired plating amount can be ensured within the time of the reheating holding. The plating time is preferably set to be, for example, 1 to 10 seconds.

There are the following three patterns of (I) to (III) as a combination of the hot-dip galvanizing treatment; and only the heating and without performing the plating treatment, in the reheating.

(I) Only the heating is carried out, and thereafter, the hot-dip galvanizing treatment is carried out.

(II) The hot-dip galvanizing treatment is carried out, and thereafter, only the heating is carried out.

(III) Only the heating is carried out, and thereafter, the hot-dip galvanizing treatment is carried out, and further, only the heating is carried out, in this order.

The reheating temperature at which only the heating is carried out and the temperature of the plating bath used for performing the hot-dip galvanizing may be different from each other. In the present invention, heating or cooling may be carried out from one temperature to the other temperature. Furnace heating, induction heating, or the like may be adopted as a method for the heating.

A high-strength hot-dip galvannealed steel sheet having a tensile strength of 980 MPa or more and being excellent in formability and crashworthiness according to the present invention can also be produced by subjecting a steel satisfying a component composition described above to hot rolling with a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being the Ar₃ point or higher to 900° C. or lower, coiling with a coiling temperature being 600° C. or lower, and cooling to room temperature; cold rolling; heating, at an average heating rate of 10° C./second or more, to a temperature region of the Ac₃ point or higher, and soaking by holding in the temperature region for 50 seconds or more; cooling at an average cooling rate of 10° C./second or more, to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and the Ms point or lower; and heating and holding in a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower for 50 seconds or more, and after performing hot-dip galvanizing within a holding time, further performing an alloying treatment and thereafter cooling to room temperature. In other words, the steps until heating to the temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower are the same as those of the above-described method for producing a high-strength cold-rolled steel sheet according to the present invention, so that the hot-dip galvanizing and the holding for 50 seconds or more that is carried out in the above temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower may be simultaneously carried out in the same step, and thereafter the hot-dip galvanized layer may be alloyed, followed by cooling down to room temperature.

The alloying treatment temperature is not particularly limited; however, when the alloying treatment temperature is too low, the alloying does not proceed sufficiently, so that the alloying treatment temperature is preferably 450° C. or higher, more preferably 460° C. or higher, and still more preferably 480° C. or higher. However, when the alloying treatment temperature is too high, the alloying proceeds too much, and the Fe concentration in the plating layer becomes high, thereby deteriorating the plating adhesion property. From such a viewpoint, the alloying treatment temperature is preferably 550° C. or lower, more preferably 540° C. or lower, and still more preferably 530° C. or lower.

The alloying treatment lime is not particularly limited and may be adjusted so that the hot-dip galvanized layer may be alloyed. The alloying treatment time is preferably, for example, 10 to 60 seconds. The alloying treatment is carried out after performing the hot-dip galvanizing treatment for a predetermined period of time within the temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower, so that the time needed for the alloying treatment is not included in the holding time within the temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower.

After performing the hot-dip galvanizing within the holding time in the temperature region of higher than the cooling slop temperature T° C. to 550° C. or lower and performing the alloying treatment in accordance with the needs, the steel sheet may be cooled down to room temperature. The average cooling rate during the cooling is not particularly limited; however, the average cooling rate is preferably, for example, 0.1° C./sec or more, more preferably 0.4° C./sec or more. Further, the average cooling rate is preferably, for example, 200° C./sec or less, more preferably 150° C./sec or less.

The high-strength cold-rolled steel sheet according to the present invention has a tensile strength of 980 MPa or more. The tensile strength is preferably 1000 MPa or more, more preferably 1010 MPa or more. Further, the above high-strength cold-rolled steel sheet is excellent in formability as evaluated by ductility and stretch-flangeability, and also is excellent in crashworthiness.

The ductility can be evaluated by strength-elongation balance. In the present invention, those in which a product of the tensile strength TS (MPa) and the elongation EL (%) is 13000 MPa·% or more are rated as acceptable. The value of TS×EL is preferably 13100 MPa·% or more, more preferably 13200 MPa·% or more.

The stretch-flangeability can be evaluated by strength-hole expansion ratio balance. In the present invention, those in which a product of the tensile strength TS (MPa) and the hole expansion ratio λ (%) is 40000 MPa·% or more are rated as acceptable. The value of TS×λ is preferably 41000 MPa·% or more, more preferably 42000 MPa·% or more.

The crashworthiness can be evaluated by strength-VDA bending angle balance. In the present invention, those in which a product of the tensile strength TS (MPa) and the VDA bending angle (°) is 90000 MPa·° or more are rated as acceptable. The value of TS×VDA bending angle is preferably 90500 MPa·° or more, more preferably 91000 MPa·° or more.

The thickness of the high-strength cold-rolled steel sheet according to the present invention is not particularly limited; however, the steel sheet is preferably a thin steel sheet having a thickness of, for example, 6 mm or less.

The present application claims the rights of priority based on Japanese Patent Application No. 2015-071437 filed on Mar. 31, 2015 and Japanese Patent Application No. 2015-225506 filed on Nov. 18, 2015. The entire contents of the specifications of Japanese Patent Application No. 2015-071437 and Japanese Patent Application No. 2015-225506 are incorporated in the present application by reference.

EXAMPLES

Hereafter, the present invention will be described more specifically by way of Examples; however, the invention is not limited by the following Examples and can be carried out while including additional modifications within a scope conforming to the gist disclosed heretofore and hereinafter, all such modifications being encompassed within the technical scope of the invention.

A steel containing the components given in the following Table 1 with the balance being iron and inevitable impurities was prepared by ingot-making and subjected to hot rolling, cold rolling, and continuous annealing to produce a cold-rolled steel sheet. In the following Table 1, “-” means that the corresponding element is not contained. The following Table 1 also show the temperature of the Ar₃ point calculated on the basis of the above formula (ii) and the temperature of the Ac₃ point calculated on the basis of the above formula (iii). Further, FIG. 1 shows one example of a heat treatment pattern that was carried out in the continuous annealing. In FIG. 1, the reference sign 1 denotes a heating step, 2 a soaking step, 3 a cooling step, 4 a reheating holding step, and 5 a cooling stop temperature.

Hot Rolling

A slab obtained by ingot-making was heated to 1250° C., and hot rolling was carried out to a sheet thickness of 2.3 mm with the rolling reduction in the final stand of finish rolling being set to be a rolling reduction shown in the following Table 2-1 or 2-2 and with the finish rolling end temperature being set to be a temperature shown in the following Table 2-1 or 2-2. After the hot rolling, the steel sheet was cooled down to a coiling temperature shown in the following Table 2-1 or 2-2 at an average cooling rate of 30° C./sec, followed by coiling. After the coiling, the steel sheet was cooled in air to room temperature, so as to produce a hot-rolled steel sheet.

Cold Rolling

After the obtained hot-rolled steel sheet was pickled to remove surface scale, cold rolling was carried out to produce a cold-rolled steel sheet having a thickness of 1.2 mm.

Continuous Annealing

The obtained cold-rolled steel sheet was subjected to continuous annealing based on the heal treatment pattern shown in FIG. 1. That is, the obtained cold-rolled steel sheet was heated as a heating step at an average heating rate shown in the following Table 2-1 or 2-2 up to the soaking temperature shown in the following Table 2-1 or 2-2, and was held at the soaking temperature as a soaking step. The following Table 2-1 or 2-2 shows the soaking time. Further, the following Table 2-1 or 2-2 shows a value calculated by subtracting the temperature of the Ac₃ point from the soaking temperature.

After the soaking, the steel sheet was cooled as a cooling step at an average cooling rate shown in the following Table 2-1 or 2-2 down to the cooling slop temperature T° C. shown in the following Table 2-1 or 2-2.

After the cooling, the steel sheet was heated to the reheating temperature shown in the following Table 2-1 or 2-2 and was held at the reheating temperature as a reheating holding step, followed by cooling down to room temperature to produce a lest sample material. The following Table 2-1 or 2-2 shows the reheating holding lime. Also, the following Table 2-1 or 2-2 shows a value calculated by subtracting the cooling slop temperature T from the reheating temperature.

Further, the Ms point was calculated in accordance with the above formula (iv) based on the component composition shown in the following Table 1. The results are shown in the following Tables 2-1 and 2-2. The following Tables 2-1 and 2-2 also show a value obtained by subtracting the temperature of the Ms point from the cooling stop temperature T.

No. 11 shown in the following Table 2-1 and No. 29 shown in the following Table 2-2 are samples in which the reheating holding step was not carried out after the cooling was stopped at the cooling stop temperature T shown in the following Table 2-1 or 2-2. That is, in No. 11, the steel sheet was cooled with the cooling stop temperature T set to be 440° C., and thereafter cooled to 350° C., which was lower than that temperature, and held at 350° C. for 600 seconds. For the sake of convenience, the following Table 2-1 gives 350° C. in the section of the reheating temperature and gives 600 seconds in the section of the reheating holding time. In No. 29, the steel sheet was cooled with the cooling stop temperature T set to be 350° C., and thereafter cooled to 330° C., which was lower than that temperature, and held at 330° C. for 300 seconds. For the sake of convenience, the following Table 2-2 gives 330° C. in the section of the reheating temperature and gives 300 seconds in the section of the reheating holding time.

Electrogalvanization

No. 15 shown in the following Table 2-1 is a sample in which the above test sample material was immersed into a galvanizing bath of 55° C. to perform an electrogalvanization treatment and thereafter washed with water and dried to produce an electrogalvanized steel sheet. The electrogalvanization treatment was carried out with an electric current density set to be 40 A/dm². The galvanizing adhesion amount was 40 g/m² per one surface. In the electrogalvanization treatment, washing treatments such as degreasing with alkaline aqueous solution immersion, washing with water, and pickling or the like were carried out as appropriate, so as to produce a test sample material having an electrogalvanized layer on the surface of the cold-rolled steel sheet. In the following Table 2-1, the section of classification for No. 15 gives “EG”.

Hot-Dip Galvanizing

No. 36 shown in the following Table 2-2 is a sample in which the above test sample material was immersed into a hot-dip galvanizing bath of 460° C. to perform a hot-dip galvanizing treatment, thereby to produce a hot-dip galvanized steel sheet. The hot-dip galvanizing adhesion amount was 30 g/m² per one surface. In the following Table 2-2, the section of classification for No. 36 gives “GI”.

Hot-Dip Galvannealing

No. 6 shown in the following Table 2-1 is a sample in which the above test sample material was immersed into a hot-dip galvanizing bath of 460° C. to perform a hot-dip galvanizing treatment, followed by heating to 500° C. to perform an alloying treatment, thereby to produce a hot-dip galvannealed steel sheet. The hot-dip galvannealing adhesion amount was 30 g/m² per one surface. In the following Table 2-1, the section of classification for No. 6 gives “GA”.

Test sample materials in which none of the electrogalvanization treatment, hot-dip galvanizing treatment, and hot-dip galvannealing treatment was carried out are denoted as “cold-rolled” in the section of classification in the following Tables 2-1 and 2-2.

With respect to the obtained test sample materials, a metal structure was observed by the following procedure.

Observation of Metal Structure Area Ratio of Ferrite and Hard Phase

After the cross-section of the obtained test sample material was polished, the test sample material was subjected to nital corrosion, followed by performing observation at the position of ¼ of the sheet thickness in three fields of view at a magnification of 1000 times with a scanning electron microscope, so as to capture a photomicrograph image. The observation field of view was such that one field of view had a size of 100 μm×100 μm. With the lattice interval set to be 5 μm, the area ratio of ferrite was measured by the point counting method with the number of lattice points being 20×20, and an average value of the three fields of view was calculated. The calculation results are shown in the following Tables 3-1 and 3-2. The area ratio of ferrite was calculated by excluding the area ratio of the hard phase that existed in the ferrite phase.

In a similar manner, a sum area ratio of pearlite and cementite was measured by the point counting method, and an average value of the three fields of view was calculated. The calculation results are shown in the following Tables 3-1 and 3-2. The sum area ratio of pearlite and cementite is denoted as “other structures” in the following Tables 3-1 and 3-2.

In the present Examples, the structure other than ferrite, pearlite, and cementite calculated by the point counting method was assumed to be a hard phase. In other words, a value obtained by subtracting the area ratio of ferrite and the sum area ratio of pearlite and cementite from 100% was calculated as an area ratio of the hard phase. The results are shown in the following Tables 3-1 and 3-2.

As a result of observation of a specific structure constituting the hard phase, it was found out that the hard phase included quenched martensite and retained γ and included at least one selected from the group consisting of bainitic ferrite, bainite, and tempered martensite.

Volume Ratio V_(γ) of Retained γ

The obtained test sample material was polished down to the position of ¼ of the sheet thickness with use of a sandpaper of #1000 to #1500, and further the surface was subjected to electrolytic polishing down to the depth of 10 to 20 μm, followed by measuring the volume ratio V_(γ) of retained γ with use of an X-ray diffractometer. Specifically, “RINT 1500” manufactured by Rigaku Corporation was used as the X-ray diffractometer and, with use of a Co target, a power of 40 kV−200 mA was output to measure the range of 40° to 130° in terms of 2θ. The volume ratio V_(γ) of retained γ was quantitated on the basis of the obtained bcc (α) diffraction peaks (110), (200), and (211) and fcc (γ) diffraction peaks (111), (200), (220), and (311). The results are shown in the following Tables 3-1 and 3-2.

Area Ratio V_(MA) and Average Circle-Equivalent Diameter of MA Structure

After the cross-section of the obtained test sample material was polished, the test sample material was subjected to LePera corrosion, followed by performing observation at the position of ¼ of the sheet thickness in three fields of view at a magnification of 1000 times with an optical microscope, so as to capture a photomicrograph image. The observation field of view was such that one field of view had a size of 100 μm×100 μm. The portion whitened by LePera corrosion was regarded as the MA structure. With the lattice interval set to be 5 μm, the area ratio of the MA structure was measured by the point counting method with the number of lattice points being 20×20, and an average value of the three fields of view was calculated. The calculation results are shown in the following Tables 3-1 and 3-2.

Upon subjecting the photomicrograph image captured with the optical microscope to image analysis, the average circle-equivalent diameter d of each MA structure was calculated, and an average value was determined. The results are shown in the following Tables 3-1 and 3-2.

Ratio of Area Ratio V_(MA) of MA Structure to Volume Ratio V_(γ) of Retained γ

The ratio V_(MA)/V_(γ) of the area ratio V_(MA) of the MA structure to the volume ratio V_(γ) of the retained γ was calculated on the basis of the volume ratio V_(γ) of the retained γ and the area ratio V_(MA) of the MA structure calculated by the above-described procedure. The calculation results are shown in the following Tables 3-1 and 3-2.

Next, with respect to the obtained test sample material, the mechanical properties, ductility, stretch-flangeability, and crashworthiness were evaluated by the following procedure.

Evaluation of Mechanical Properties and Ductility

A No. 5 test piece defined in JIS Z2201 was cut out so that the direction perpendicular to the rolling direction of the obtained test sample material would be a longitudinal direction. With use of this test piece, a tensile test was carried out so as to measure the tensile strength TS and the elongation EL. The measurement results are shown in the following Tables 3-1 and 3-2.

In the present Examples, the samples in which the tensile strength was 980 MPa or more were evaluated as having a high strength and being acceptable, whereas the samples in which the tensile strength was less than 980 MPa were evaluated as having an insufficient strength and being a reject.

Also, the value of tensile strength TS×elongation EL was calculated on the basis of the measured values of tensile strength TS and elongation EL. The calculation results are shown in the following Tables 3-1 and 3-2. The value of TS×EL indicates a strength-elongation balance and serves as an index for evaluating the ductility.

In the present Examples, the samples in which the value of TS×EL was 13000 MPa·% or more were evaluated as having an excellent ductility and being acceptable, whereas the samples in which the value of TS×EL was less than 13000 MPa·% were evaluated as having a poor ductility and being a reject.

Evaluation of Stretch-Flangeability

In order to evaluate the stretch-flangeability of the test sample material, a hole expansion lest was carried out according to the Japan Iron and Steel Federation Standard JFS T 1001, so as to measure the hole expansion ratio λ. The measurement results are shown in the following Tables 3-1 and 3-2.

Also, the value of tensile strength TS×hole expansion ratio λ was calculated on the basis of the measured values of tensile strength TS and hole expansion ratio λ. The calculation results are shown in the following Tables 3-1 and 3-2. The value of TS×λ indicates a strength-hole expansion ratio balance and serves as an index for evaluating the stretch-flangeability.

In the present Examples, the samples in which the value of TS×λwas 40000 MPa·% or more were evaluated as having an excellent stretch-flangeability and being acceptable, whereas the samples in which the value of TS×λ was less than 40000 MPa·% were evaluated as having a poor stretch-flangeability and being a reject.

Evaluation of Crashworthiness

It is disclosed in the following literature that the crashworthiness is correlated to a bending angle.

Literature: P. Larour, H. Pauli, T. Kurz, T. Hebesberger. “Influence of post uniform tensile and bending properties on the crash behavior of AHSS and press-hardening steel grades”, IDDRG2010

Accordingly, a bending test was carried out under the following conditions on the basis of the VDA standard (VDA238-100) defined by the German Association of the Automotive Industry. The displacement at the maximum load measured by the bending test was converted into an angle according to the VDA standard, so as to determine the bending angle. The conversion results are shown in the following Tables 3-1 and 3-2.

Measurement Conditions

Test method: support with rolls, pressing-in of punch

Roll diameter: φ30 mm

Punch shape: tip end R=0.4 mm

Distance between rolls: 2.9 mm

Punch pressing-in speed: 20 mm/min

Test piece dimension: 60 mm×60 mm

Bending direction: direction perpendicular to the rolling direction

Testing machine: SIMAZU AUTOGRAPH 20 kN

Also, the value of tensile strength TS×VDA bending angle° was calculated on the basis of the values of the tensile strength TS measured in the tensile lest and the VDA bending angle. The calculation results are shown in the following Tables 3-1 and 3-2.

In the present Examples, the samples in which the value of TS×VDA was 90000 MPa·° or more were evaluated as having an excellent crashworthiness and being acceptable, whereas the samples in which the value of TS×VDA was less than 90000 MPa·° were evaluated as having a poor crashworthiness and being a reject.

On the basis of the above results, samples satisfying ail of the requirements: the value of TS being 980 MPa or more, the value of TS×EL being 13000 MPa·% or more, the value of TS ×λbeing 40000 MPa·% or more, and the value of TS×VDA being 90000 MPa·° or more were regarded as the present invention examples and listed as being acceptable in the total evaluation section of the following Tables 3-1 and 3-2. On the other hand, samples in which one or more of the value of TS, the value of TS×EL, the value of TS×λ. and the value of TS×VDA failed to satisfy the above acceptance standard were regarded as the comparative examples and listed as being a reject in the total evaluation section of the following Tables 3-1 and 3-2.

TABLE 1 Steel Component (mass %) type C Si Mn P S Al Cr Mo Ti Nb V Cu A 0.19 1.53 2.38 0.02 0.002 0.02 — — — — — — B 0.23 2.55 2.18 0.04 0.001 0.03 — — — — — — C 0.16 1.56 2.09 0.02 0.001 0.03 — — — — — — D 0.25 2.25 2.34 0.05 0.002 0.02 0.1 — — — — — E 0.18 2.39 1.85 0.02 0.001 0.02 — 0.2 — — — — F 0.29 1.97 2.34 0.04 0.001 0.01 — — 0.08 — — — G 0.41 2.35 2.00 0.04 0.001 0.03 — — — 0.07 — — H 0.12 1.76 2.22 0.05 0.001 0.03 — — — — 0.10 — I 0.13 2.01 2.29 0.01 0.002 0.01 — — — — — 0.10 J 0.20 1.07 2.30 0.02 0.002 0.02 — — — — — — K 0.24 1.37 2.40 0.03 0.003 0.01 — — — — — — L 0.19 2.73 2.13 0.01 0.002 0.03 — — — — — — M 0.22 2.89 2.00 0.02 0.001 0.01 — — — — — — N 0.18 2.14 1.55 0.01 0.003 0.03 — — — — — — O 0.20 2.25 1.72 0.01 0.001 0.03 — — — — — — P 0.21 2.32 2.89 0.05 0.001 0.02 — — — — — — Q 0.16 1.83 4.67 0.01 0.003 0.01 — — — — — — R 0.24 1.89 6.22 0.03 0.002 0.02 — — — — — — S 0.07 1.59 2.57 0.03 0.003 0.03 — — — — — — T 0.17 0.58 2.50 0.02 0.002 0.01 — — — — — — U 0.17 2.15 1.18 0.03 0.002 0.01 — — — — — — Ar₃ Ac₃ Steel Component (mass %) point point type Ni B Ca Mg REM N O (° C.) (° C.) A — — — — — 0.003 0.002 660 840 B — — — — — 0.004 0.001 664 901 C — — — — — 0.005 0.001 694 862 D — — — — — 0.004 0.001 644 881 E — — — — — 0.003 0.002 690 903 F — — — — — 0.002 0.001 634 883 G — — — — — 0.002 0.002 622 865 H — — — — — 0.003 0.001 697 911 I 0.10 — — — — 0.002 0.001 680 866 J — 0.0024 — — — 0.005 0.001 664 820 K — — 0.0015 — — 0.004 0.002 643 824 L — — — 0.0019 — 0.005 0.001 681 899 M — — — — 0.0030 0.003 0.002 682 902 N — — — — — 0.005 0.002 731 893 O — — — — — 0.003 0.001 709 887 P — — — — — 0.002 0.001 613 877 Q — — — — — 0.002 0.002 488 783 R — — — — — 0.002 0.002 339 738 S — — — — — 0.004 0.002 684 885 T — — — — — 0.005 0.001 659 796 U — — — — — 0.002 0.001 762 912

TABLE 2 Annealing step Hot rolling step Reheating holding Final Heating Soaking Cooling Reheating Finish rolling stand Average Soaking Average Cooling stop temperature- Reheating end rolling Coiling heating Soaking temperature- Soaking cooling Cooling stop Ms temperature T- Reheating cooling stop holding Steel temperature rate temperature rate temperature Ac₃ point time rate temperature T point Ms point temperature temperature T time No. type (° C.) (%) (° C.) (° C./sec) (° C.) (° C.) (sec) (° C./sec) (° C.) (° C.) (° C.) (° C.) (° C.) (sec) Classification 1 A 880 15 500 15 870 30 300 15 190 391 −201 300 110 600 Cold-rolled 2 A 880 15 500 15 870 30 300 15 25 391 −366 400 375 600 Cold-rolled 3 A 880 10 550 2 910 70 550 10 350 391 −41 420 70 600 Cold-rolled 4 A 880 10 550 15 910 70 300 10 420 391 29 450 30 600 Cold-rolled 5 B 850 15 550 10 910 9 300 15 280 379 −99 380 100 600 Cold-rolled 6 B 850 15 550 10 910 9 300 15 250 379 −129 440 190 300 GA 7 B 1000 15 550 10 910 9 300 15 330 379 −49 440 110 600 Cold-rolled 8 B 880 15 700 10 910 9 300 15 360 379 −19 420 60 600 Cold-rolled 9 B 880 15 550 10 910 9 300 1 360 379 −19 420 60 600 Cold-rolled 10 C 880 15 550 15 880 18 400 15 370 417 −47 420 50 600 Cold-rolled 11 C 880 15 550 15 880 18 400 15 440 417 23 350 −90 600 Cold-rolled 12 D 880 15 550 10 910 29 300 15 220 364 −144 350 130 600 Cold-rolled 13 D 880 35 550 10 910 29 300 15 300 364 −64 430 130 600 Cold-rolled 14 D 880 3 550 10 910 29 300 15 350 364 −14 460 110 600 Cold-rolled 15 E 880 7 500 10 910 7 300 10 300 409 −109 440 140 600 EG 16 E 880 7 500 10 840 −63 300 10 300 409 −109 440 140 600 Cold-rolled 17 F 880 20 550 15 900 17 300 15 200 347 −147 300 100 600 Cold-rolled 18 G 880 20 550 15 880 15 300 15 180 300 −120 250 70 600 Cold-rolled 19 H 880 15 550 15 920 9 300 15 300 433 −133 400 100 600 Cold-rolled 20 I 880 15 550 15 910 44 300 15 250 423 −173 350 100 600 Cold-rolled 21 J 880 15 550 15 850 30 300 391 −141 330 330 600 Cold-rolled 22 K 880 10 550 15 880 56 300 20 200 367 −167 220 20 600 Cold-rolled 23 K 880 10 550 15 880 56 300 20 350 367 −17 500 150 5 Cold-rolled 24 K 880 15 550 15 880 56 300 20 350 367 −17 650 300 1000 Cold-rolled 25 L 880 15 500 15 910 11 300 20 200 401 −201 250 50 600 Cold-rolled 26 M 880 15 500 15 930 28 300 20 250 392 −142 300 50 600 Cold-rolled 27 N 880 15 450 15 910 17 300 20 250 426 −176 300 50 600 Cold-rolled 28 O 880 15 450 15 900 13 300 20 250 408 −158 350 100 600 Cold-rolled 29 O 880 30 450 15 900 13 300 15 350 408 −58 330 −20 300 Cold-rolled 30 P 880 15 550 15 900 23 300 15 250 356 −116 400 150 600 Cold-rolled 31 Q 880 15 550 15 850 67 300 10 300 333 −33 500 200 1000 Cold-rolled 32 R 880 15 550 15 850 112 300 10 200 244 −44 500 300 1000 Cold-rolled 33 S 880 15 550 15 900 15 300 10 300 445 −145 400 100 600 Cold-rolled 34 T 880 15 550 15 880 84 300 10 250 400 −150 300 50 600 Cold-rolled 35 U 880 15 550 15 930 18 300 10 400 441 −41 500 100 600 Cold-rolled 36 A 880 15 500 15 870 30 550 30 250 391 −141 420 170 600 GI 37 P 880 15 550 15 900 23 300 15 350 366 −16 450 100 300 Cold-rolled 38 C 880 15 600 7 910 48 450 10 400 417 −17 450 50 300 Cold-rolled 39 A 880 15 500 15 850 10 300 7 370 391 −21 430 60 200 Cold-rolled 40 B 850 15 550 15 910 9 300 15 140 379 −239 180 40 600 Cold-rolled 41 N 880 15 550 15 910 17 300 20 70 426 −356 380 310 600 Cold-rolled 42 C 880 15 550 15 880 18 300 15 250 417 −167 370 120 100 Cold-rolled 43 B 900 15 500 15 910 9 100 20 230 379 −149 400 170 600 Cold-rolled

TABLE 3 Structure fraction Average MA circle-equivalent Hard Other Retained Y structure diameter of MA Ferrite phase structures V_(Y) V_(MA) structure No. (area %) (area %) (area %) (vol %) (area %) (μm) V_(MA)/V_(Y) 1 1 95 4 6 7 1.0 1.17 2 2 95 3 3 1 0.7 0.33 3 5 91 4 10 12 2.2 1.20 4 4 94 2 11 15 2.7 1.36 5 3 94 3 10 11 1.2 1.10 6 3 94 3 11 14 1.4 1.27 7 4 93 3 12 17 2.3 1.42 8 3 92 5 14 19 2.4 1.36 9 28 65 7 16 21 1.8 1.31 10 3 94 3 10 13 1.1 1.30 11 3 95 2 8 15 1.7 1.88 12 3 94 3 7 9 1.2 1.29 13 6 90 4 10 12 2.5 1.20 14 4 94 2 11 15 2.2 1.36 15 3 95 2 11 13 1.3 1.18 16 32 65 3 14 19 1.5 1.36 17 2 96 2 11 14 1.4 1.27 18 2 96 2 13 15 1.7 1.15 19 1 97 2 7 8 1.2 1.14 20 3 93 4 8 9 1.1 1.13 21 2 97 1 7 8 1.4 1.14 22 1 97 2 5 6 1.0 1.20 23 1 97 2 14 53 4.3 3.79 24 2 82 16 2 2 0.9 1.00 25 2 94 4 6 9 1.2 1.13 26 5 93 2 9 10 1.4 1.11 27 6 91 3 7 8 1.3 1.14 28 4 94 2 8 9 1.3 1.13 29 3 95 2 6 11 2.3 1.83 30 1 97 2 8 9 1.2 1.13 31 0 98 2 6 8 1.6 1.33 32 0 97 3 7 8 0.9 1.14 33 2 96 2 4 4 1.4 1.00 34 0 97 3 2 3 1.0 1.50 35 18 74 8 10 12 1.8 1.20 36 3 94 3 8 11 1.4 1.38 37 5 93 2 21 24 1.7 1.14 38 5 93 2 13 18 2.2 1.38 39 23 74 3 8 11 1.9 1.38 40 3 95 2 6 5 0.9 0.83 41 3 95 2 4 3 1.0 0.75 42 6 92 2 6 4 0.8 0.67 43 4 92 4 8 10 1.0 1.25 Material properties TS EL λ VDA TS × EL TS × λ TS × VDA Total No. (MPa) (%) (%) (°) (MPa · %) (MPa · %) (MPa · °) evaluation 1 1306 11 52 75 14366 67912 97950 Acceptable 2 1421 6 39 68 8526 55419 96628 Reject 3 1042 14 34 91 14588 35428 94822 Reject 4 993 15 32 83 14895 31776 82419 Reject 5 1321 12 38 72 15852 50196 95112 Acceptable 6 1125 15 42 88 16875 47250 93375 Acceptable 7 1295 12 26 70 15540 33670 90650 Reject 8 1226 12 24 74 14712 29424 90724 Reject 9 1104 19 17 84 20976 18768 92736 Reject 10 1021 15 61 104 15315 62281 106184 Acceptable 11 1012 14 51 93 14168 51612 83996 Reject 12 1423 10 32 66 14230 45536 93918 Acceptable 13 1287 11 25 65 14157 32175 83655 Reject 14 1154 18 29 79 15002 33466 91166 Reject 15 1056 15 51 89 15840 53856 93984 Acceptable 16 991 23 24 92 22793 23784 91172 Reject 17 1352 12 81 70 16224 41912 94640 Acceptable 18 1546 9 28 60 13914 48288 92760 Acceptable 19 1032 14 52 91 14448 53664 93912 Acceptable 20 1153 13 42 82 14989 48426 94546 Acceptable 21 1232 12 40 80 14784 49280 98560 Acceptable 22 1510 10 31 63 15100 46810 95130 Acceptable 23 1642 5 8 31 8210 13136 50902 Reject 24 846 11 19 79 9306 16074 66834 Reject 25 1373 11 32 68 15108 43936 93364 Acceptable 26 1298 11 37 71 14278 48026 92158 Acceptable 27 1193 13 41 78 15509 48913 93054 Acceptable 28 1104 14 46 84 15456 50784 92736 Acceptable 29 1337 11 23 58 14707 30751 77546 Reject 30 1125 13 45 88 14625 50625 93375 Acceptable 31 1218 12 38 79 14616 46284 96222 Acceptable 32 1339 10 32 69 13390 42848 92391 Acceptable 33 1092 10 55 88 10920 60060 96096 Reject 34 1274 7 42 72 8918 53508 91728 Reject 35 991 15 29 95 14865 26739 94145 Reject 36 1108 15 41 92 16545 45223 101476 Acceptable 37 1004 15 42 95 15060 42168 95380 Acceptable 38 991 16 39 94 15356 38649 93154 Reject 39 1162 13 15 79 15106 17430 91798 Reject 40 1536 10 31 62 15360 47616 95232 Acceptable 41 1052 11 68 87 11572 71536 91524 Reject 42 1294 11 54 71 14234 69876 91874 Acceptable 43 1253 13 42 77 16289 52626 96481 Acceptable

From Tables 1, 2-1, 2-2, 3-1, and 3-2, the following considerations can be made.

Tables 3-1 and 3-2, all of the samples rated as “acceptable” in the total evaluation section are steel sheets satisfying the requirements defined in the present invention, and all of the value of TS×EL, the value of TS×λ, and the value of TS×VDA determined in accordance with the tensile strength TS satisfy the acceptance standard values. It will be understood that these steel sheets have good formability as evaluated by ductility and stretch-flangeability, and are excellent in stretch-flangeability in particular, and also in crashworthiness.

In contrast, the samples rated as “reject” in the total evaluation section are steel sheets that do not satisfy one or more of the requirements defined in the present invention, and at least one of ductility, stretch-flangeability. and crashworthiness could not be improved. The details are as follows.

No. 2 is a sample in which a predetermined amount of retained γ and the MA structure could not be ensured because the cooling stop temperature T after the soaking was an extremely low temperature of 25° C. which was lower than 100° C., so that the value of V_(MA)/V_(γ) was below the defined range. As a result, the value of TS×EL was small, so that the ductility could not be improved.

Nos. 3 and 38 are samples in which the MA structure was coarsened because the average heating rate after the coiling was too small. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved.

No. 4 is a sample in which the MA structure was coarsened because the cooling stop temperature T after the soaking was too high and exceeded the temperature region of 100° C. or higher and the Ms point or lower. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved. Also, the value of TS×VDA was small, so that the crashworthiness could not be improved.

No. 7 is a sample in which the MA structure was coarsened because the finish rolling end temperature was too high. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved.

No. 8 is a sample in which the MA structure was coarsened because the coiling temperature was too high. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved.

Nos. 9 and 39 are samples in which fertile was excessively generated because the average cooling rate after the soaking was too small. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved.

No. 11 is a sample in which the value of V_(MA)/V_(γ) was too large because the cooling stop temperature T after the soaking was too high and exceeded the temperature region of 100° C. or higher and the Ms point or lower and because the reheating holding was not carried out after the cooling. As a result, the value of TS×VDA was small, so that the crashworthiness could not be improved.

No. 13 is a sample in which the MA structure was coarsened because the rolling reduction at the final stand during the finish rolling was loo high and exceeded the range defined in the present invention. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved. Also, the value of TS×VDA was small, so that the crashworthiness could not be improved.

No. 14 is a sample in which the MA structure was coarsened because the rolling reduction at the final stand during the finish rolling was too low and was below the range defined in the present invention. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved.

No. 16 is a sample in which ferrite was excessively generated because the soaking was carried out al a temperature below the Ac₃ point. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved.

No. 23 is a sample in which the MA structure was coarsened because the reheating holding time was too short As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved. Further, the MA structure was generated excessively. As a result, the value of TS×EL was small, so that the ductility could not be improved. Also, the value of V_(MA)/V_(γ) was too large. As a result, the value of TS×VDA was small, so that the crashworthiness was deteriorated.

No. 24 is a sample in which decomposition of austenite occurred and a predetermined amount of retained γ and the MA structure could not be ensured because the reheating temperature carried out after the cooling was too high. As a result, TS was small.

No. 29 is a sample in which the MA structure was coarsened and the value of V_(MA)/V_(γ) was too large because the rolling reduction at the final stand during the finish rolling was too high and exceeded the range defined in the present invention and because the reheating holding was not carried out after the cooling. As a result, the value of TS×λ was small, so that the stretch-flangeability could not be improved. Further, the value of TS×VDA was small, so that the crashworthiness could not be improved.

No. 33 is a sample in which the C amount was too small, so that a retained γ amount within the range defined in the present invention could not be ensured. As a result, the value of TS×EL was small, so that the ductility was deteriorated.

No. 34 is a sample in which the Si amount was too small, so that a retained γ amount within the range defined in the present invention could not be ensured. As a result, the value of TS×EL was small, so that the ductility was deteriorated.

No. 35 is a sample in which the Mn amount was too small, so that the hardenability was insufficient, and ferrite was excessively generated. As a result, the value of TS×λ was small, so that the stretch-flangeability was deteriorated.

No. 41 is a sample in which a predetermined amount of retained γ could not be ensured because the cooling stop temperature T after the soaking was below 100° C. As a result, the value of TS×EL was small, so that the ductility could not be improved.

REFERENCE SIGNS

1 Healing step

2 Soaking step

3 Cooling step

4 Reheating holding step

5 Cooling stop temperature 

1. A cold-rolled steel sheet having a tensile strength of 980 MPa or more, the cold-rolled steel sheet comprising, in mass %: C: 0.10% or more to 0.5% or less, Si: 1.0% or more to 3% or less, Mn: 1.5% or more to 7% or less, P: more than 0% to 0.1% or less, S: more than 0% to 0.05% or less, Al: 0.005% or more to 1% or less, N: more than 0% to 0.01% or less, and O: more than 0% to 0.01% or less, wherein a metal structure at a position of ¼ of a sheet thickness satisfies (1) to (4) below: (1) when the metal structure is observed with a scanning electron microscope, an area ratio of ferrite relative to a whole of the metal structure is 0% or more to 10% or less, with a balance being a hard phase including quenched martensite and retained austenite and including at least one selected from the group consisting of bainitic ferrite, bainite, and tempered martensite, (2) when the metal structure is measured by X-ray diffractometry, a volume ratio V_(γ) of retained austenite relative to the whole of the metal structure is 5% or more to 30% or less, (3) when the metal structure is observed with an optical microscope, an area ratio V_(MA) of an MA structure, in which quenched martensite and retained austenite are combined, relative to the whole of the metal structure is 3% or more to 25% or less, and an average circle-equivalent diameter of the MA structure is 2.0 μm or less, and (4) a ratio V_(MA)/V_(γ) of the area ratio V_(MA) of the MA structure to the volume ratio V_(γ) of the retained austenite satisfies a formula (i) below: 0.50≦V _(MA) /V _(γ)≦1.50   (i).
 2. The cold-rolled steel sheet according to claim 1, further comprising, as other elements, one or more of any of (a) to (e) below, in mass %: (a) at least one selected from the group consisting of Cr: more than 0% to 1% or less and Mo: more than 0% to 1% or less, (b) at least one selected from the group consisting of Ti: more than 0% to 0.15% or less, Nb: more than 0% to 0.15% or less, and V: more than 0% to 0.15% or less, (c) at least one selected from the group consisting of Cu: more than 0% to 1% or less and Ni: more than 0% to 1% or less, (d) B: more than 0% to 0.005% or less, and (e) at least one selected from the group consisting of Ca: more than 0% to 0.01% or less, Mg: more than 0% to 0.01% or less, and REM: more than 0% to 0.01% or less.
 3. An electrogalvanized steel sheet having an electrogalvanized layer on a surface of the high-strength cold-rolled steel sheet according to claim
 1. 4. A hot-dip galvanized steel sheet having a hot-dip galvanized layer on a surface of the cold-rolled steel sheet according to claim
 1. 5. A hot-dip galvannealed steel sheet having a hot-dip galvannealed layer on a surface of the cold-rolled steel sheet according to claim
 1. 6. A method for producing a cold-rolled steel sheet according to claim 1, having a tensile strength of 980 MPa or more, the method comprising: hot rolling steel with a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being an Ar₃ point or higher to 900° C. or lower, coiling the steel with a coiling temperature being 600° C. or lower, and cooling the steel to room temperature; cold rolling the steel; heating the steel, at an average heating rate of 10° C./second or more, to a temperature region of an Ac₃ point or higher, and soaking the steel while holding the steel in the temperature region for 50 seconds or more; cooling the steel at an average cooling rate of 10° C./second or more, to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and an Ms point or lower; and heating and holding the steel in a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower for 50 seconds or more, and thereafter cooling the steel to room temperature.
 7. A method for producing a hot-dip steel sheet according to claim 1, having a tensile strength of 980 MPa or more and being excellent in formability and crashworthiness, the method comprising: hot rolling steel with a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being an Ar₃ point or higher to 900° C. or lower, coiling the steel with a coiling temperature being 600° C. or lower, and cooling the steel to room temperature; cold rolling the steel; heating the steel, at an average heating rate of 10° C./second or more, to a temperature region of an Ac₃ point or higher, and soaking the steel while holding the steel in the temperature region for 50 seconds or more; cooling the steel at an average cooling rate of 10° C./second or more, to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and an Ms point or lower; and heating and holding the steel in a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower for 50 seconds or more, and after performing hot-dip galvanizing within a holding time, cooling the steel to room temperature.
 8. A method for producing a hot-dip steel sheet according to claim 1, having a tensile strength of 980 MPa or more and being excellent in formability and crashworthiness, the method comprising: hot rolling steel with a rolling rate at a final stand of finish rolling being 5 to 25% and with a finish rolling end temperature being an Ar₃ point or higher to 900° C. or lower, coiling the steel with a coiling temperature being 600° C. or lower, and cooling the steel to room temperature cold rolling the steel; heating the steel, at an average heating rate of 10° C./second or more, to a temperature region of an Ac₃ point or higher, and soaking the steel while holding the steel in the temperature region for 50 seconds or more; cooling the steel at an average cooling rate of 10° C./second or more, to an arbitrary cooling stop temperature T° C. that lies in a temperature range of 100° C. or higher and an Ms point or lower; and heating and holding the steel in a temperature region of higher than the cooling stop temperature T° C. to 550° C. or lower for 50 seconds or more, and after performing hot-dip galvanizing within a holding time, further performing an alloying treatment and thereafter cooling the steel to room temperature. 